U.S. patent number 5,704,355 [Application Number 08/492,998] was granted by the patent office on 1998-01-06 for non-invasive system for breast cancer detection.
Invention is credited to Jack E. Bridges.
United States Patent |
5,704,355 |
Bridges |
January 6, 1998 |
Non-invasive system for breast cancer detection
Abstract
A system for detecting an incipient tumor in living tissue such
as that of a human breast in accordance with differences in
relative dielectric characteristics. A generator produces a
non-ionizing electromagnetic input wave of preselected frequency,
usually exceeding three gigahertz, and that input wave is used to
illuminate the living tissue, being effectively focused into a
small, discrete volume within the tissue to develop a non-ionizing
electromagnetic wave at that position. The illumination location is
moved over a portion of the living tissue in a predetermined
scanning pattern. Scattered signal returns collected from the
living tissue are collected to develop a scattered return signal.
The scattered return signal is employed to detect any anomaly,
caused by differences in relative dielectric characteristics, that
is indicative of the presence of a tumor in the scanned living
tissue.
Inventors: |
Bridges; Jack E. (Park Ridge,
IL) |
Family
ID: |
26953839 |
Appl.
No.: |
08/492,998 |
Filed: |
June 21, 1995 |
Related U.S. Patent Documents
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Application
Number |
Filing Date |
Patent Number |
Issue Date |
|
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269691 |
Jul 1, 1994 |
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Current U.S.
Class: |
600/407; 607/101;
607/154 |
Current CPC
Class: |
A61B
5/05 (20130101); A61B 5/0507 (20130101); A61B
5/4312 (20130101); A61B 6/0435 (20130101); A61B
6/502 (20130101) |
Current International
Class: |
A61B
5/05 (20060101); A61B 6/00 (20060101); A61B
005/05 () |
Field of
Search: |
;128/653.1,633,664,665,660.01,660.02,660.06,915 ;364/413.25 ;600/2
;606/2,12,33 ;250/330-334,358.1,363.01 ;607/100,101,97,154 |
References Cited
[Referenced By]
U.S. Patent Documents
Primary Examiner: Casler; Brian L.
Attorney, Agent or Firm: Dorn, McEachran, Jambor &
Keating
Parent Case Text
This application is a continuation-in-part of U.S. Ser. No.
08/269,691, filed Jul. 1, 1994 now abandoned.
Claims
I claim:
1. A non-invasive system utilizing non-ionizing electromagnetic
millimeter waves of minimal thermal heating capacity for detection
of a tumor in a breast, comprising:
a generator for generating a non-ionizing high-frequency
electromagnetic input wave;
illumination means for creating an effectively focussed
non-ionizing electromagnetic beam from the input wave and directing
said beam to impinge upon an effective focal point at a
predetermined position within a breast;
wave impedance matching means, in the illumination means, matching
the impedance of the illumination means to the wave impedance of
normal breast tissue;
a wave guide for applying the input wave from the generator to the
breast through the illumination means;
focal point shifting means, connected to the illumination means,
for shifting the effective focal point across the breast in a
predetermined pattern to scan selected incremental volumes within
the breast;
at least one scattered wave collector positioned to intercept
scattered waves from the incremental volumes within the breast and
develop a return signal representative of the scattered waves from
within the breast;
and a receiver, including a detector, connected to the scattered
wave collector, for detecting anomalies in the return signal to
identify a tumor and its location in the breast.
2. A non-invasive system for detection of a tumor in a breast
according to claim 1 and further comprising:
separator means, connected to the scattered wave collector, for
separating the scattered wave signals from the input wave in
developing the return signal.
3. A non-invasive system for detection of a tumor in a breast
according to claim 2 in which the separator means includes a
circulator.
4. A non-invasive system for detection of a tumor in a breast
according to claim 2 in which the separator means includes
polarization-responsive means for separating the input wave from
the return signal based on polarization of the return signal.
5. A non-invasive system for detection of a tumor in a breast
according to claim 2 in which:
the separator means includes a pulse source of repetitive pulse
signals; and
the system further comprises display means, connected to the pulse
source of the separator means and to the receiver, for displaying
the returns as a function of time;
the rise time for each pulse signal being no greater than 300
pico-seconds.
6. A non-invasive system for detection of a tumor in a breast
according to claim 2 in which the pulse source is a part of a
frequency-modulated pulse compression system that employs a
frequency bandwidth of at least two gigahertz.
7. A non-invasive system for detection of a tumor in a breast
according to claim 2 and further comprising compensation means for
compensating for change in the dielectric constant of the breast as
a function of frequency.
8. A non-invasive system for detection of a tumor in a breast,
according to claim 2, in which a synthetic time-domain response is
developed from the Fourier inversion of the complex input impedance
data as the frequency of the illumination signal is progressively
changed over a bandwidth of at least two gigahertz.
9. A non-invasive system for the detection of a tumor, according to
claim 8, and further comprising means to compensate for the changes
in the equipment behavior as a function of frequency.
10. A non-invasive system for the detection of a tumor, according
to claim 8, and further comprising means to compensate for the path
loss attenuation as the illuminating signal progresses into the
breast.
11. A non-invasive system for detection of a tumor in a breast
according to claim 1, in which:
the reflection receiver is a part of the illumination means;
and further comprising separator means, connected to the scattered
wave collector, for separating the scattered wave signals from the
input wave in developing the return signal.
12. A non-invasive system for detection of a tumor in a breast
according to claim 1 in which:
the illumination means comprises a globular antenna filled with a
first dielectric medium;
the illumination means further comprises a connecting device,
connecting the antenna to the breast, filled with a second
dielectric medium; and
the dielectric constants of the breast, the first dielectric
medium, and the second dielectric medium are all approximately
equal to each other.
13. A non-invasive system for detection of a tumor in a breast
according to claim 12 in which the globular antenna is of truncated
ellipsoidal configuration and functions as a part of the
transmitter and a part of the collector.
14. A non-invasive system for detection of a tumor in a breast,
according to claim 12, in which the dielectric constants are in a
range of four to twenty.
15. A non-invasive system for detection of a tumor in a breast
according to claim 1 in which the focal point shifting means
includes a mechanical scanner to change the location of the
illuminator means relative to the breast.
16. A non-invasive system for detection of a tumor in a breast
according to claim 15 and further comprising:
focal point indication means, connected to the mechanical scanner;
and
imaging means, connected to the receiver and to the focal point
indication means, for displaying an image of the breast including a
representation of any tumor therein.
17. A non-invasive system for detection of a tumor in a breast
according to claim 1 in which the connection from the generator to
the receiver includes a phase shift circuit for shifting the input
wave, as applied to one of the detectors, by an odd multiple of
90.degree. relative to the input wave as supplied to the other
detector.
18. A non-invasive system for detection of a tumor in a breast
according to claim 17 in which each of the detectors is a hybrid
tee.
19. A non-invasive system for detection of a tumor in a breast
according to claim 1 in which the distance from the effective focal
point to the effective aperture of the illuminator is no greater
than four times the diameter of the effective aperture.
20. A non-invasive system for detection of a tumor in a breast,
according to claim 1, comprising at least two scattered wave
collectors, disposed on opposite sides of the breast.
21. A non-invasive system for detection of a tumor in a breast,
according to claim 1, in which the receiver includes a directional
coupler.
22. An illumination means for a non-invasive system for the
detection of a tumor in a breast according to claim 1
comprising:
an array of a plurality of independently excitable wave guides,
each having an excitation end and an open end;
means to note the position of the contact point of each illuminator
wave guide between the open end of the wave guide and the surface
of the breast, with no more than a minimum space between the wave
guide and the breast;
means to control the phase angle of the input wave of each
illuminator wave guide at its contact point in accordance with the
position of the contact point; and
means to change the phase angle of the input wave of each
illuminator wave guide at its contact point such that the
individual waves that propagate from each of the illuminator wave
guides into the breast add constructively at an effective focal
point within a predetermined incremental volume within the
breast.
23. An illumination means for a non-invasive system for detection
of a breast tumor according to claim 22 and further comprising
means to move the array of wave guides and the interface
mechanically to scan the breast.
24. An illumination means according to claim 22 and further
comprising:
means to controllably and independently position the open ends of
the illuminator wave guides into predetermined positions on the
surface of the breast.
25. An illumination means according to claim 22 in which the
illuminator wave guides are each filled with materials that have
dielectric characteristics similar to that for the human
breast.
26. A scattered wave collector for a non-invasive system for the
detection of a tumor in the breast, including an illumination means
according to claim 22, that further includes a scattered wave
collector positioned to intercept waves scattered from the
effective focal point, comprising:
an array of a plurality of collector wave guides, each having an
open end;
means to note the position of the contact point of the open end of
each collector wave guide and the surface of the breast; and
means to control the phase angle of each of the waves collected by
each collector wave guide such that the collected scattered waves
that propagate from the effective focal point in the breast to each
of the collector wave guides on the surface of the breast are
constructively combined.
27. A wave collection means for a non-invasive system for the
detection of a tumor, according to claim 26, in which the
illuminator wave guides are also the collector wave guides.
Description
BACKGROUND OF THE INVENTION
Breast cancer is one of the leading causes of death for women.
About one out of eight or nine women are expected to develop tumors
of the breast, and about one out of sixteen to twenty are expected
to die prematurely from breast cancer.
Mammography or other X-ray methods are currently most used for
detection of breast cancers. However, every time a mammogram is
taken, the patient incurs a small risk of having a breast tumor
induced by the ionizing radiation properties of the X-rays used
during the mammogram. Also, the process is costly and sometimes
imprecise. Accordingly, the National Cancer Institute has not
recommended mammograms for women under fifty years of age, who are
not as likely to develop breast cancers as are older women.
However, while only about twenty two percent of breast cancers
occur in women under fifty, data suggests that breast cancer is
more aggressive in pre-menopausal women. Furthermore, women under
forty are getting the disease in increasing numbers--about eleven
thousand annually now--and no one knows why.
Mammograms require interpretation by radiologists. One radiologist
has said "I generally can spot cancers between five and ten
millimeters in diameter. The prognosis is excellent then." However,
about ten to fifteen percent of tumors of this size are not
detected. One study showed major clinical disagreements for about
one-third of the same mammograms that were interpreted by a group
of radiologists. Further, many women find that undergoing a
mammogram is a decidedly painful experience.
Thus, alternative methods to detect breast cancers are needed,
especially those that do not entail added risks, that can detect
tumors as small as two millimeters in diameter, that are not unduly
unpleasant to the patient, and that can be used for mass screening.
A screening system is needed because extensive studies have
demonstrated that early detection of small breast tumors leads to
the most effective treatment. While X-ray mammography can detect
lesions of approximately five mm or larger, the accuracy may range
between 30% and 75%, depending on the skill of the diagnostic
radiologist. Repeated X-ray examinations, however, are not
encouraged because these may become carcinogenic. These
considerations, in addition to cost considerations, have led
physicians to recommend that women wait until the age of fifty
before having routine mammograms. One solution would be a
non-ionizing, non-invasive, and low cost detection or screening
method. It could greatly increase without hazard the number of
patients examined and would identify those patients who need
diagnostic X-ray examinations, where the added hazards and costs
could be justified. Thus, there is a need for a low-cost,
non-invasive, screening method.
About one in eight women develop breast cancers and about one in
sixteen die prematurely from this disease. Despite strong
encouragement, less than half of the millions of women who should
be are routinely screened. Some of the reasons are cost and
discomfort experienced during mammography. Other concerns are the
additional risks associated with ionizing radiation, especially for
routine exams for women under fifty. However, while only twenty two
percent of breast cancers occur in women under fifty, data suggest
that breast cancer is more aggressive in pre-menopausal women. A
screening procedure need only identify breasts with abnormalities.
The precision and imaging requirements associated with diagnostic
purposes and treatment monitoring, while desirable, need not
apply.
There are several generic detection methods: sonic, chemical,
nuclear and non-ionizing electromagnetic. The sonic, chemical and
nuclear (such as MRI) techniques have been under study for some
time and, while some interesting approaches are being followed,
none have been publicized as being available in the near future for
low cost screening.
Non-ionizing electromagnetic methods have also been under
investigation. Studies have considered the use of electromagnetic,
non-ionizing methods to detect or image portions of the human body.
An excellent summary of such activity is presented in a publication
entitled "Medical Applications of Microwave Imaging", edited by L.
E. Larsen and J. H. Jacobi, IEEE Press 1986.* These activities
include microwave thermography, radar techniques to image
biological tissues, microwave holography and tomography, video
pulse radar, frequency modulation pulse compression techniques for
biological imaging, microwave imaging with diffraction tomography,
inverse scattering approaches, and medical imaging using an
electrical impedance. The publications in this book contain about
five hundred citations, some of which are duplicates. The
technology cited not only includes electromagnetic disciplines, but
also notes related studies in sonic imaging and seismic imaging. To
update these data, the IEEE transactions on Medical Imaging,
Biomedical Engineering, Microwave Theory and Techniques and
Antennas and Propagation have been reviewed. Also surveyed was the
publication Microwave Power and Engineering. This update has
indicated little significant progress in the aforementioned
electromagnetic techniques that would be important to detect
Many important reasons exist for this lack of progress. In the case
of microwave thermography, adequate depth of penetration, along
with the required resolution, may not be realized, except for large
cancers. In the case of holography, reflections at the skin-air
interface tend to mask the desired returns from breast tumors
beneath the skin. Further, illuminating the entire volume of a
breast either requires excessive power (with possible biological
hazards) or acceptance of poor signal-to-noise ratios. In the case
of through-the-body electromagnetic techniques, such as tomography,
the attenuation characteristics of the body are such that long
wavelengths are usually used, with an attendant loss of resolution.
Imaging by determining perturbations in body impedance caused by
the presence of tumors as sensed by multi-electrode arrays have
been either inadequate in sensitivity or subject to false
alarms.
A millimeter wave FM radar weapons detection system developed and
tested for the FAA (DTFA03-87-C-00056) by the inventor employed a
94 GHz FM radar operating with a 300 Mhz bandwidth. A half-meter
diameter antenna with a half inch spot size focused the radiated 94
GHz energy through the air onto a possible passenger boarding an
aircraft. This system successfully detected both metallic and
plastic weapons, with an overall detection probability of 96.2%.
The false alarm rate was 31.09%. It was hoped, initially, that the
system could be used to detect breast cancers, since there was some
empirical evidence suggested that the 94 GHz waves were penetrating
the skin sufficiently that some portions of the shoulder blades
could be resolved. However, subsequent research has disclosed that
the air-skin interface would not only enlarge the spot size, but
would reflect a very substantial fraction of the impinging
waveform.
To mitigate the resolution problem, a much higher frequency is
needed to realize a usable spot size. However, the use of higher
frequencies greatly increases the path attenuation of the
penetrating energy, thereby introducing major design difficulties.
These findings largely negated the use of this system for breast
cancer detection. Nevertheless, the results of this FAA project
suggested that at least some features of a millimeter wave weapons
detection system, designed from existing data, could be revised and
integrated into a successful prototype system for detecting breast
tumors.
SUMMARY OF THE INVENTION
The objective of this invention is to provide a system to propagate
non-ionizing electromagnetic waves having wavelengths not much
greater than three times the circumference of the smallest tumor to
be detected, preferably having wavelengths, in normal breast
tissue, of the order of thirty millimeters or less and preferably
of the order of ten millimeters. Propagation is effected without
incurring intractable path losses, while at the same time being
able to discern breast tumors of the order of three millimeters.
The penetration is realized by: 1) avoiding interface reflections
by employing media that have about the same dielectric constant as
the breast tissues; 2) choosing a frequency (and wavelength) that
readily penetrates normal breast tissue; and 3) providing means to
extract tumor-scattered power from the applied or impinging power.
The desired resolution is achieved by: 1) choosing a frequency such
that its wavelength in breast tissue is comparable to the minimum
size tumor to be detected; 2) using a wide aperture antenna that
focuses the mmw energy at discrete points within the breast; and 3)
relying on significant differences between the dielectric
properties of the normal breast tissue and those of the breast
tumors. Optimum operation is usually achieved at frequencies in the
range of three to ninety gigahertz.
A principal feature of this invention includes means to introduce
microwave or millimeter wave energy into a breast with a minimum of
interface reflections and loss of resolution (or increased spot
size). This is done by means of dielectric materials in the
illuminator that have about the same relative dielectric constant
as the breast tissue and by use of gels, liquids, slurries and/or
solids that have a similar relative dielectric constant around the
breast to further suppress interface gaps that could cause
reflections and loss of resolution.
Another important feature is the selection of a band of operating
frequencies wherein the attenuation of the propagating energy in a
non-lactating breast is relatively small, preferably of the order
of 1.5 to 15 dB/cm, in combination with an antenna or illuminator
aperture size that produces a spot size preferably in a range of
about 2.5 to 12 millimeters in normal, non-lactating breast
tissue.
Another important feature comprises the use of a wide aperture
scanning system. The construction of the scanner is such that the
focus of the energy introduced is scanned at different depths, at
depth increments comparable to the depth of focus, to provide a
quasi-three-dimensional picture of the backscattered returns. To
overcome path anomalies that might cause ambiguous results,
different scanning patterns can be employed to average out such
effects. Also, advantage can be taken of other features inherent in
electromagnetic propagation systems, such as the use of different
polarization effects, including circular polarization, and
enhancement of the backscatter cross-section wherein the
circumference of the tumor is equal to the wavelength. Also, use of
forward and side scatter can be employed to help resolve
ambiguities.
Yet another important feature employs techniques that aid in
separating the desired scattered returns from a tumor from those
originating either directly from the impinging waveform or from
spurious reflections from scatterers of no interest. This may be
done by "passive methods", such as employed in microwave circuits
(magic tees or circulators) or by tumor-unique scattering phenomena
(wherein the polarization, side-scatter, forward-scatter returns or
tumorinduced resonant effects are utilized). Additionally, "active
methods", such as time-gating or pulse-compression methods
(sometimes employed in modern radar systems) may also be used.
Another feature of this invention is the use of a stepped frequency
technique to develop a synthetic time domain response. As opposed
to applying a large amplitude short duration pulse and then using
time-gating or the use of swept frequency FM "Chirp" radar pulse
compression methods, the stepped or swept frequency input impedance
method can be more easily implemented. The dwell time at each
frequency can be adjusted to give adequate signal-to-noise ratios,
digital processing and control can be used, and the hardware needed
to implement this method is available.
Another feature of this invention is the use of confocal
techniques, where the focal point of the illumination and the focal
point of the collection system are nearly the same point in the
breast tissue. Such arrangements suppress the effects of incidental
sources of scattering that might occur at locations outside the
common focal point.
Another feature is the combined use of the confocal method with the
stepped frequency synthetic time domain method, especially for
detecting anomalies at depth. On one hand, the confocal method is
most effective at shallow depths, and loses its ability to suppress
incidental scattering for deeper tumors. The synthetic time domain
method, if used separately from the confocal arrangement with more
commonly available antennas, will generate back scatter from
sources over a wide area. Scatter from such incidental sources
could mask the desired returns from any tumor. However, the
combined use will provide more benefit than would be suggested by
the performance of each subsystem separately. The confocal method
suppresses clutter sources (incidental scattering) that are
transverse to the direction of propagation and the time domain
system suppresses clutter sources in the longitudinal
direction.
Another feature of the invention is convenience to conduct
screening. As opposed to other microwave methods that require
access to nearly all sides of the breast, the method noted here
needs access to only one side.
Another feature of the invention is that it can provide
non-hazardous screening functions, such that breasts, over time,
can be compared to detect abnormalities that would not otherwise be
possible with an ionizing approach or more expensive methods, such
as MRI.
One version of the invention includes a quasi holographic technique
wherein the amplitude and phase of the scattered returns are
compared to a reference signal and subsequently used to form some
type of three dimensional display. A modified interferometer
technique can be used to do this. The interferometer provides 3-D
displays of the backscattered power and the cumulative phase shift
of the returns with respect to a reference point.
BRIEF DESCRIPTION OF THE DRAWINGS
The following figures are used to explain the concepts and design
of the breast cancer detection system of the invention:
FIG. 1A, is a conceptual view an active millimeter wave breast
cancer detection system, with a patient;
FIG. 1B illustrates displays for plural focal lengths, with the
generalized system of FIG. 1A;
FIG. 2 is a simplified block diagram that illustrates the principal
functions of a mmw breast cancer detection system constructed in
accordance with the invention;
FIG. 3 is a graph of relative dielectric constants of muscle, fat,
breast tissue and breast cancer as reported by various
investigators;
FIG. 4 is a graph of conductivity of muscle, fat, breast tissue and
breast cancers as reported by various investigators;
FIG. 5 is a graph of attenuation, wavelength, and depth of
penetration in normal breast tissue as a function of frequency,
based on the data presented in FIGS. 3 and 4;
FIG. 6 is a block diagram of a mmw breast cancer detection system,
according to the invention, that employs a "passive" signal
separation technique in combination with a conventional heterodyne
receiver to detect tumor-scattered returns;
FIG. 7 is a block diagram of a breast cancer detection system,
again according to the invention, that employs phase coherent
detection;
FIG. 8 is a diagram of resolution (or spot size) and depth of focus
as functions of the diameter of an aperture or lens and of
wavelength;
FIG. 9 shows Snell's Law effects that illustrate quasi-optical
propagation from a medium with a low relative dielectric constant
into a medium with a very high relative dielectric constant;
FIG. 10 is a schematic cross-sectional illustration of a large
aperture illuminator in the form of an ellipsoidal reflector in
combination with a boot that contains a material having relative
dielectric properties similar to those for normal breast
tissues;
FIG. 11 is a graph that shows the backscatter cross-section of a
perfectly conducting sphere normalized to the cross sectional area
of the sphere as a function of the circumference-to-wavelength
ratio;
FIG. 12 presents a simplified block diagram of another detection
system, according to the invention, that employs an "active" or
time domain technique to help extract power scattered by a tumor
from applied or impinging mmw power;
FIG. 13 illustrates an array of double ridged wave guides that can
be used to replace the ellipsoidal reflector;
FIG. 14 presents a simplified functional block diagram on how the
phased array can be controlled to position the focal point without
the need for mechanical scanning;
FIG. 15 shows how the a wave guide like that of FIG. 13 can be
positioned directly on the breast for screening purposes; and
FIG. 16 illustrates how forward scattering can be sensed by a
confocal arrangement wherein the focal point of the receiving array
tracks the focal point of the illuminating array.
DESCRIPTION OF THE PREFERRED EMBODIMENTS
The use of electromagnetic microwave or millimeter waves offers
several advantages over x-ray mammography in detecting incipient
breast cancers. (To simplify this discussion both microwave and
millimeter wavelength regimes will be referred to as mm waves, or
mmw.) Non-ionizing electromagnetic systems can be operated at
sufficiently low levels so as to preclude biological hazards. A
contrast ratio of the order of 20:1 is potentially usable for mm
waves in tissue, whereas there is less than a few per cent range of
densities for X-rays for soft tissue. The tissue-mm wave
interaction also 5 exhibits additional phenomena that can be drawn
upon to enhance the performance. For example, when the diameter of
a highly conducting sphere (e.g., an incipient cancer) is of the
order of a wavelength in the breast tissue, a resonance effect
occurs that increases the effective scattering cross-section of the
tumor. If the tumor is non-spherical, then the polarization of the
scattered waves may be different than that of the impinging
waveform. In some cases, side-scattered or forward scattered energy
can also be utilized. For purposes of this specification, tissue-mm
waves are defined in terms of wavelength in a medium having a
dielectric constant like that of breast tissue, not air. Thus, the
operating frequency for an electromagnetic wave source used in the
inventive system is preferably in the range of three to ninety
GHz.
Other than the use of millimeter wave and microwave thermography to
detect breast cancers, there has been little activity toward use of
such mm wave approaches to detect breast cancers. As noted earlier,
some of the problems that have to be overcome are formidable.
First, simply flooding the torso of a female with mmw energy
introduces numerous problems. How does one single out the scattered
return from a three millimeter circumference tumor out of the
immensely larger scattered returns from the torso? How is the
defocusing effect of the air-skin interface overcome? Is the breast
tissue sufficiently transparent, at mmw frequencies, to propagate
energy into and out of the breast? Are the dielectric properties of
the tumors sufficiently different from normal breast tissue for
effective detection of small (e.g., three mm circumference)
incipient cancers?
To understand the invention and its novel features, the basic
concept will first be briefly described. Next, the ability of the
millimeter wave electromagnetic energy to penetrate normal breast
tissues will be demonstrated. Then, the special equipment and
operating conditions will be described to realize the needed high
resolution simultaneously with good penetration.
FIGS. 1A and lB illustrate the basic concepts. FIG. 1A illustrates,
on a conceptual basis, possible prototype equipment. The patient 21
arranges one of her breasts 22 to contact an illuminator 23 as
shown. Mm waves are generated within the equipment housing 24.
These mm waves are then propagated into the selected breast 22 as a
refracted or reflected electromagnetic mm wave that is focused at a
predetermined point or volume (voxel) within the breast. This is
done by means of a unique combination of an interface and focusing
apparatus, as described hereinafter. Further apparatus is used to
cause the focal point of the beam to scan different small volumes
or voxels within the breast. When this happens, the scattered mmw
energy from any tumor present in the breast becomes much larger
that other scattering sources, since the dielectric properties of a
tumor are radically different than that of the breast tissue. The
scattered returns may be collected as backscattered power via the
same interface and focusing apparatus that is used to propagate the
mmw power into the breast. The collected power can then be
processed by either analog or digital methods to form an image of
the tumor.
A stepped FM sweep similar to pulse compression in "Chirp" radar to
synthesize a time domain response to isolate shallow from in-depth
scattering can be used to mitigate the effects of heterogeneity in
the dielectric characteristic of the breast. The functional goal of
the combined confocal and time-domain features is to isolate the
returns from tumors from spurious returns generated by
heterogeneity in adjacent normal tissues.
Electromagnetic waves in the mm wave region, in combination with
the shape and dielectric properties of tumors in the breast, offer
additional methods to detect the presence of a tumor beyond using
just simple back, forward, or side scatter. In some cases, the
tumor can exhibit both internal and external electromagnetic
resonances which are unique to its presence. Such resonances can be
detected by varying the mmw frequency, by observing changes in
polarization, by observing transient responses to an impulse
function, or by noting changes in the ratio of the forward, side,
backscattered and spurious returns. If the geometry of the tumor is
asymmetrical, then the plane of polarization of the scattered
energy may change; this change can be used to confirm the presence
of a small tumor.
The amount of collected backscattered energy and its accumulated
phase shift (or time of flight or round trip time delay) can be
presented in a 3-D format, as shown generally in FIG. 1B. For
illustrative purposes, it is assumed that the impinging energy can
be selectively and sharply focused into three vertical planes that
are parallel to the patient's chest, wherein the x-y planes at
maximum depth 25, medium depth 26, and shallow depth 27 are shown.
The three coordinates show the backscatter returns 28, the "x"
coordinate 30 and the "y" coordinate 29. Small vertical lines 31
are shown for numerous combinations of x and y coordinates.
The amplitudes or heights of most of these lines 31 are
proportional to the non-target returns that can arise from, for
example, the tissues that surround the rib cage. Note that a very
large return 32 exists in the center of the medium depth display
26. This large return 32 is assumed to arise from a tumor that is
at the focus of the impinging energy in the medium depth plane 26.
In the center of the Shallow plane 27 there is a somewhat smaller
response 33 caused by the tumor intercepting and only scattering a
small portion of the impinging beam. Note that in the center of the
deeper plane 25, the return 34 is smaller because, it is assumed,
the focused energy has largely been scattered by the tumor in the
medium depth plane 26 before it arrives at the center of the deeper
plane 25.
FIG. 2 presents a block diagram that illustrates the principal
functions of the mmw breast cancer detection and imaging apparatus.
Microwave or millimeter wave power is generated by a mmw power
generator 41. This power is supplied to a power and signal director
43 via a cable or waveguide 42. The power output 44 from the
director 43 flows to an illuminator 47 via a waveguide 46. The
illuminator 47, via a scanning plate 49 of dielectric material,
causes the power to be focused at a point 62 within the breast 22.
A scan control 48, via a mechanical connection 50, causes the
illuminator 47 to move along the plate 49 in a predetermined
scanning pattern. When the focus of the power encounters a tumor
61, backscattered power 45 is collected by illuminator 47 and is
returned, via waveguide 46, to the power and signal director
43.
To prevent the applied power from swamping or masking returns from
the tumor 61, means must be included to extract the desired return
or signal from the tumor from the applied power. The initial
function of the director 43 is to direct the mmw power output 44
from the generator 41 to the focusing illuminator 47 through the
cable or waveguide 46. The director 43 also is employed to extract
the tumor-scattered returns 45 that are collected by the focusing
illuminator 47. The extracted returns 45 from the power and signal
director 43 are applied to a mmw receiver 53 via a cable or
waveguide 52.
The requisite directing action of the director 43 can be realized
by several "passive" means, such as a balanced bridge circuit or
magic tee, a directional coupler, or a circulator (see Ramo et al.
(1965) Fields and Waves in Communication Electronics, John Wiley
and Sons, New York, sections 11.17, 11.8 and 9.16). "Active" means
of separating the applied power 44 from the tumor-scattered power
45 are possible in the time domain. For example, very short
duration pulses of mmw energy can be applied and the returns
separated by time gating methods. Other "active" methods currently
employed in some modern radar systems can be used, such as pulse
compression, chirp or frequency modulation radar; see Skolnik,
Introduction to Modern Radar Systems, McGraw-Hill (1980).
The focusing illuminator 47 of FIG. 2 has several functions. One
principal function is to focus the applied power at a predetermined
point within the breast 22. Another principal function is to
condition the spatial distribution of dielectric material to
enhance resolution. Yet another function is to suppress dielectric
and electrical interface reflections that could mask the scattered
returns from a possible tumor 61 in the breast 22 of the patient
21. These functions may be done by matching the wave propagation
characteristic or dielectric constant of the illuminator 47 and the
scanning plate 49 to that of the breast 22 and also matching the
electrical interface between the cable/waveguide 46 and the
focusing illuminator 47 by means of electrical matching networks,
such as the mmw equivalent of a "pi" or "tee" or "L" network.
The scan control 48 controls the position of the focal point 62 of
the illuminator 47 via a mechanical connection 50 that slides the
illuminator 47 over the scanning plate 49 in a predetermined
scanning pattern. This action provides x and y positioning of the
focal point. Alternatively, other techniques may be used in
conjunction with the scan control 48 to create an apparent focal
point, such as by means of phased arrays or synthetic aperture
methods.
The scattered returns 45 from a possible tumor or other scattering
sources are applied to the mmw receiver 53 via the wave guide 52
and the power and signal director 43. This mmw receiver 53 may be a
conventional heterodyne receiver that provides an output
proportional to the power received. Alternatively, using a
waveguide 58 connected from the mmw generator 41 to the receiver
53, a reference signal can be compared with the return signal 45 to
develop composite phase and amplitude data.
The outputs from the mmw receiver 53 are supplied, via a cable 54,
to a signal processing and display unit 55. This unit 55, with a
further input from the scan control 48 via a cable 51, processes
the received data into a suitable display, such as illustrated in
FIG. 1B.
In the case of screening for breast cancer, the performance
requirements can be relaxed, since the detection of an abnormality
is the real goal. This can be done by comparing the returns from
one breast with the other. In addition, year-to-year examination
data can be compared. As shown in FIG. 2, information via cable
bundle 70 on the returns from each breast can be compared; see
block 71. Cable bundle 72 carries similar data for storage and
subsequent comparison via block 73 after each yearly
examination.
Various known comparison techniques can be used for this purpose.
For example, a transparency of a positive image taken of the breast
at one time may be overlain with a transparency of a negative image
taken at a later time. Any significant return on the positive is
presented as a very light gray area in the refrence-gray background
and the return taken a later time is displayed as a dark area in
the reference-gray background. If no change has occurred, the light
gray area on the positive and the dark gray area on the negative
will tend to cancel and result in a nearly reference-gray density.
If some change has occurred in a specific area, the images will not
cancel in this region, and the abnormality will be indicated as
either a darker or lighter region in the reference-gray background.
A similar process can be done digitally, and the difference
displayed visually in a two dimensional display for a given "slice"
or depth into the breast.
FIGS. 3, 4 and 5 provide data that demonstrate that non-lactating
breast tissue has different dielectric properties than either
tumors or muscle tissues. Moreover, the attenuation of mm waves in
such breast tissue is not excessive in the 5 to 15 GHz region and
hence permits reasonable operating conditions for "passive" power
and signal directors. Additional attenuation can be tolerated by
the use of "active" power and signal directors such that operation
up to sixty GHz is possible.
FIG. 3 summarizes data on relative permittivity, scale 101, as a
function of frequency, scale 102. These data demonstrate that the
relative dielectric properties of low-water-content tissues and
normal breast tissues are significantly lower than for
high-water-content tissues and tumors, either human or non-human.
The low-water content data for curve 103 were developed by
Chaudhary (1984) for human breast tumors. Johnson (1972) developed
the data for curve 105 for fat, bone and low-water content tissue.
Edrich (1976) generated the data for cattle fat, shown in the curve
107. Burdette (1986) generated in vivo data for canine fat,
illustrated in a curve 109. The high-water-content data for another
curve 104 was developed by Chaudhary (1984) for human breast
tumors. Johnson (1972) developed data for muscle and high water
content tissues, shown in a curve 106. Rogers (1983) generated the
data, shown in a curve 108, for mouse tumors. Edrich (1986)
collected data for canine muscle, illustrated in a curve 110.
Burdette (1986) provided in vivo data, shown in curve 112, for
canine muscle tissue. Note that in the case of muscle or tumor
tissues, the relative dielectric constant is of the order of forty
or more, depending on the frequency. In the case of
low-water-content tissues, such as breast or fat, the dielectric
constant is in the order of five to ten, as measured for in vitro
studies. The in vivo measurements of Burdette (1986), shown in
curves 109 and 112, show an approximate increase by a factor of two
in the relative permittivity over the data developed by Johnson
(1972), curves 105 and 106. The in vitro breast tissue measurements
by Chaudhary (1984), curves 103 and 104, fall somewhat in between
the in vitro values developed by Johnson (1972) and the in vivo
measurements of Burdette (1986).
FIG. 4 presents similar data on the conductivity of both low and
high-water-content tissues. The conductivity in mhos/meter, scale
121, is the ordinate and the frequency, curve 122, is the abscissa.
The low-water-content tissues are human breast tissues, shown in a
curve 123 derived from Chaudhary (1984). The low-water-content fat
and bone of the curve 125 is from Johnson (1972). Cattle fat, shown
in a curve 127 is from Edrich (1986). The high-water-content
tissues of the curve 124 are human breast tumors, data by Chaudhary
(1984). High-water-content muscle tissue is in a curve 126, data by
Johnson (1972). Mouse tumors, shown in a curve 128, are from Rogers
(1983). Rat muscle data for a curve 130 is derived from Edrich
(1986). Canine fat data are presented in a curve 131 from Burdette
(1980), and canine muscle data in a curve 132 taken from Burdette
1980). Note that conductivity, as a function of frequency, tends to
increase substantially above 6 GHz and that the 40 to 90 GHz
measurements of Edrich (curves 127 and 130) tend to fall in line
with the trends established by measurement made up to 10 GHz.
Based on the data presented in FIGS. 3 and 4, FIG. 5 shows the
depth of penetration 140, wavelength 142, and attenuation 144 as a
function of frequency 146 for the propagation of millimeter waves
in non-lactating breast tissue. Above ten GHz, some uncertainty
associated with the trend extrapolation is suggested by the range
of possible values of the penetration depth 140 or attenuation 144.
A value of nine was used for the relative dielectric constant and
the extrapolated values of Chaudhary (relative to the data
developed by Johnson) from FIG. 4 were used for the conductivity.
From these data, it is seen that the breast tissue behaves as a
lossy dielectric for frequencies substantially exceeding five GHz,
wherein .omega.=2.pi.F and .di-elect cons.=.di-elect cons..sub.O
.di-elect cons..sub.r (permittivity of free space).times.(relative
dielectric constant), .sigma. is the conductivity, .mu. is the
permeability, f is the frequency, .lambda. is the wavelength, and
.delta. is the depth of penetration (see Ramo (1965) page 334 Sec.
6.05).
Since .omega..di-elect cons.>>.sigma., the approximate lossy
dielectric equations are as follows:
This defines the generic feasibility of the system to be described
hereinafter. There are two requirements that must be met. First,
the total path loss attenuation (in and out) should be
substantially less than the dynamic range, typically in the order
of 100 dB, wherein the dynamic range is defined in dB as equal to:
10 log[(largest signal power)/(smallest detectable signal power)].
Second, the wavelength in the irradiation apparatus (illuminator
47) and in the breast of the patient should be sufficiently small
so that small tumors can be resolved. This, for the system
discussed here, requires that, preferably, the wavelength in
illuminator 47 and in the breast tissue should not exceed two or
three times the circumference of the smallest tumor. If an
operating frequency of 15 GHz is chosen for a passive power and
signal detector, it is seen that the path loss is about 5 dB/cm, or
50 dB total path loss, in and out, for a 5 cm path length. The
wavelength at 15 GHz is about 0.6 cm, which is about equal to the
diameter of the smaller tumors.
FIG. 6 illustrates a functional block diagram of a microwave breast
cancer detection and imaging system 200 that employs a conventional
heterodyne receiver. System 200 comprises the following subsystems:
a millimeter power generator subsystem 241, a passive power and
signal director 243, a focusing illuminator subsystem 228, a
heterodyne receiver 253 employed for signal detection, a scanner
control 248, and a signal processing and display subsystem 255.
Electromagnetic wave energy flows, via the power and signal
director 243, from the power generation subsystem 241 to the
illuminator subsystem 228. The illuminator subsystem 228 comprises
three major parts: a beam focusing apparatus 247, a matching
network 226, and a dielectric equalizing interface 249. The
focusing apparatus 247 of the illuminator 228 focuses the energy
into a small point 262 within the breast of the patient 259. The
scanner 248, through a mechanical connection 250, controls the
location of the focal point 262 in three dimensions (3-D) such that
the focal point 262 is progressively positioned into each voxel
(smallest volume element) of the breast under consideration. When
the focal point encounters a tumor 261, the scattered returns are
substantially increased, since the electrical permeability and
conductivity of the tumor is greater than similar parameters for
breast tissue. The scattered returns are collected by the
illuminator 247 of subsystem 228 and then the scattered power
(arrow 245) is supplied via the matching network 226 and the power
and signal director 243 to the detection subsystem 253.
The scattered power 245 is separated from the impinging power 244
(supplied to the illuminator) by means of a circulator 224 within
the power and signal director 243. A discussion of each of the
aforementioned subsystems follows.
The power generation and control subsystem 241 is comprised of two
functional blocks: an electromagnetic wave power source 220
connected via a cable 221 to an isolator and power splitter 222.
This, in turn, is connected, via a cable 242, to the power input
port 225 of the circulator 224 in the power and signal director
243. The power output and backscattered input port 227 of the
circulator 224 is connected, via a cable 246, to the matching
network 226 at the input of the illuminator subsystem 228. The
output port 234 of the circulator 224 is connected to the signal
processor subsystem via a cable 252.
Many of the functions of these components are obvious. The
isolator/power splitter 222 electrically isolates the power source
220 from any load variations that might be introduced by the
circulator 224, the matching network 226, or other components of
the illuminator subsystem 228. The function of the circulator 224
is to extract the backscattered returns from the applied power.
Otherwise, the high level of the power applied to the illuminator
subsystem 228 would tend to mask the desired scattered returns.
Thus, the electromagnetic input signal injected into port 225 is
directed out of port 227 and thence to the matching network 226.
The backscattered returns (from the matching network 226) that are
applied to port 227 appear at port 234, wherein the amplitude of
the applied power is greatly suppressed. The purpose of the
matching network 226 in subsystem 228 is to suppress reflections
that might take place at the interfaces of different dielectric
materials or where some wave impedance discontinuity occurs in the
illuminator subsystem 228.
The performance requirements for the signal detection system 253
are not too stringent. The simplest version may use a simple
heterodyne receiver as an RF voltmeter to measure the output of the
circulator 224 at port 234. A reference signal from the power
generation subsystem 241 can be supplied to the hetrodyne receiver
253 via a conductor 258 to stabilize the local oscillators in the
receiver.
Other versions of the invention, such as the system 300 shown in
FIG. 7, offer additional signal processing options. The system 300
of FIG. 7 illustrates the use of two synchronous receivers or
detectors in a modification of the system of FIG. 6 in which only
the signal detection subsystem is changed, with subsystem 253 of
FIG. 6 replaced by a dual subsystem 353 that includes two hybrid
tee synchroneous detectors 361 and 362. The power splitter 222
(FIG. 6) provides a reference signal, on conductor 258 (FIG. 7) to
system 353 as well as to the power and signal director 243. Each of
the hybrid tee devices 361 and 362 forms a product between the
applied input signal and the composite backscattered returns.
However, one of the reference waveforms is shifted ninety degrees
with respect to the other reference waveform; the following
relationships result, where:
.omega. is the angular frequency of the millimeter waves;
.theta. is an arbitrary reference fixed phase angle;
.lambda. is the wavelength;
.chi. is the path length from the scatterer to the hybrid tee;
.beta. is the propagation phase constant and
.beta.=2.pi./.lambda.;
.chi..beta. is the accumulated phase shift.
The output from each of the hybrid tees 361,362 is the product of
the returned, scattered waveform and the reference waveform.
Considering just the low frequency components of such products, the
output of each of the hybrid tees is as follows:
The outputs can be defined as an in phase "I" vector component and
a quadrature or "Q" vector component. These are combined as vectors
so the phase angle of the combined vector becomes tan=.sup.1
(2.chi..beta.). Typically, when no tumor is at the focal point 262
(FIG. 6), the backscatter from the chest tissue-lung interface can
be assumed to form the zero reference distance for .chi.. During
scanning, the focal point may begin to encounter a tumor that is
spaced a few or more millimeter wavelengths away from the chest
muscles. When this happens, the effective distance .chi.
progressively decreases, thereby causing the equivalent phase angle
to rotate counter-clockwise. The number of rotations can be counted
to develop the total accumulated phase angle change. The above
relationships can be manipulated to present an accumulated path
delay presentation that is responsive to the approximate distance
of the scatterer from the illuminator. Such an option can be
valuable in confirming the presence of a weak scatterer and can
provide confirming location data for a strong scatter.
The dual receiver system depicted in FIG. 7 draws the reference
waveforms from the isolator-power splitter 222 via cable 258. An
attenuator-power splitter 339 is used to reduce the amplitude of
the waveform presented to the two phase shifters 340 and 341 via
appropriate cables or other conductors 352 and 351. The output
waveform of phase shifter 341 is advanced or retarded ninety
degrees relative to phase shifter 340 to provide the desired
quadrature relationship. The quadrature reference waveforms from
circuits 340 and 341 are applied, via cables 342 and 343, to the
hybrid tees 362 and 361, respectively. The output of port 234 of
the circulator 224 supplies the power from the backscattered
returns, via cable 252, to the power splitter-isolator 335. This
circuit 335 diverts the return signal equally into cables 336 and
337, thus supplying the backscattered signals to the hybrid tees
361 and 362. These tees 361 and 362 each form a product between the
reference waveform (from conductors 343 and 342, respectively) and
the backscattered signals (on lines 336 and 337, respectively). The
low frequency output from these two devices 361 and 362, on cables
345 and 346, provides critical inputs to the signal processor and
display subsystem 255 (FIG. 6). Other variations of the above
technique may be used to improve the signal-to-noise ratio, such as
modulating the reference waveforms with another frequency well
above the highest frequency of interest in the detected
backscattered return. This removes the output signal well away from
the troublesome shot noise that occurs at very low frequencies.
The scanner control subsystems 48 and 248 (FIGS. 2 and control how
the breast of the patient is scanned. In the case of the prototype
system of FIG. 2, scanner control 48 controls the x and the y
positions of an ellipsoidal reflecting antenna 47, which may be the
antenna 170 shown in FIG. 10. Several antennas of different focal
lengths may be used to access the location of a tumor. The scanner
control (48 or 248) is mechanically connected to the illuminator
(47 or 247) and to the signal processing unit (55 or 255) in each
of the described systems of FIGS. 2 and 6. Phased arrays (not
shown) could be used instead of a mechanically positioned
illuminator to realize approximately the same scanning performance.
Other methods, particularly techniques that synthesize large
aperture antennas, could also be used.
In any of the described systems the signal processing and display
subsystem (e.g., subsystem 255 in FIG. 6) can employ any number of
processing or display methods so as to suitably display the scatter
returns. It should be noted that since the scatter waveforms are
referenced to the initial unperturbed electromagnetic wave
illumination, quasi-holographic processing techniques can be
considered.
FIG. 8 defines the parameters needed to determine the spot size,
including the diameter of the aperture D, the focal distance R, the
spot diameter d, and the wavelength .lambda. of the millimeter wave
in the media. See Kay (1966) and Smith (1966) for more complete
development of relationships. Here, the spot size becomes:
As was noted earlier in regard to FIG. 5, reasonable penetration
losses of about five dB/cm occur for wavelengths of the order of
six mm. Thus, if tumors in the order of three mm in circumference
are to be resolved, the beam width or spot size should not exceed
the tumor circumference by much more than a factor of three.
Preferably, for improved spatial resolution, the wavelength should
not exceed the tumor circumference by a factor of three. To achieve
a spot diameter of 6 mm, the ratio of the focal distance R to the
aperture diameter, D should be about 0.5.
Another design consideration is the depth of field .DELTA., as
related to the aforementioned parameters and the apparent angle of
resolution .PHI.. Thus the depth of field becomes:
Again, to obtain good spatial discrimination, the focal distance R
should be small compared to the aperture diameter D.
However, short focal lengths cannot be easily developed if the
dielectric constant between the media that form an interface are
greatly different. This would be the case if an attempt is made to
propagate millimeter wave power in air and thence into the breast.
As seen in FIG. 3, the dielectric constant of breast tissue is of
the order of nine, and such a large value (relative to a value of
one for air) causes substantial reflection of the incident power at
the air-breast interface. More importantly, the apparent R/D ratio
is reduced; that can lead to a radical increase in the spot size.
This is best seen by referring to FIG. 9 (see Ramo (1965) p. 358
Sec. 6.13 for more complete background). Here the incident ray 151
impinges on a dielectric interface 150. This produces a reflected
wave 153 and a penetrating wave 155. The angle of incidence 157
must equal the angle of reflection 159. Also, Snell's Law must be
satisfied where angle 161 is the angle of the transmitted
penetrating wave 155 with respect to a normal to the plane of
incidence 150 and .di-elect cons..sub.1 and .di-elect cons..sub.2
are the dielectric constants for air and for the breast tissue,
respectively:
This interface reduction in the angle 161 of the transmitted
penetration wave 155 will tend to increase the apparent R/D ratio
(focal distance to aperture size ratio). For example, assume that a
focused mm wave front with an R/D ratio of 0.5 in air impinges on a
dielectric interface where the ratio of the relative dielectric
constant of the second media to the first media is nine. Based on
Snell's Law, the maximum value of angle 161 can be no more than
about fourteen degrees. This would increase the apparent focal
distance from R to about 4R and increase the spot diameter d by a
factor of four.
FIG. 10 illustrates one way the defocusing and reflecting effect of
the dielectric interfaces between a breast (or other tissue) and
air can be mitigated. The mm wave power from a feed point 171 in a
medium 175 is introduced, via an interface medium 176, into the
breast 177, with the respective relative dielectric constants
.di-elect cons..sub.1, .di-elect cons..sub.2 and .di-elect
cons..sub.3 made approximately the same. For illustrative purposes,
an elliptical reflector 170 is chosen; reflector 170 has an R/D
ratio of about 0.5 that would produce a spot size comparable to the
wavelength, which is of the order of 6 mm. This elliptical
reflector 170 and related apparatus is designed to exhibit two
focal points: one at the feed point 171 and the other at a point
172 in a voxel within the breast 177. An interface boot 180 is used
to contain a liquid or slurry 176 having a dielectric constant,
.di-elect cons..sub.2, that is contained by a boot wall 181, a
thin, liquid-impermeable brassiere 182, and a thin, solid
dielectric sheet 183 that has the same relative dielectric constant
as .di-elect cons..sub.1. For orientation purposes, the dash curve
178 represents the curve of the ellipse of reflector 170 if it were
to extend into the human body.
The thin brassiere 182 is caused to fit as closely as possible to
the breast 177 of the person under examination, as by withdrawing
air from the voids 179. The breast is compressed into a relatively
flat surface by the dielectric plate 183. This permits moving the
focal point 172 by moving the elliptical reflector 170 along the
surface of the dielectric plate 183 to scan the breast. The focal
point 172 may be moved upwardly by increasing the thickness of the
dielectric plate 183.
This arrangement assures that the mmw power that is applied to the
breast is focused in the voxels of interest. Future, the millimeter
wave power that is scattered from a possible tumor at the focal
point 172 returns to point 171 via paths that have equal time
delay, thus allowing constructive recombination of the scattered
returns at the feed point 171. On the other hand, power that is not
intercepted by a tumor at focal point 172 progresses on to the
breast-lung interface 185 via plural paths such as the path 186. A
portion 187 of the unscattered wave 186 progresses into the muscle
and rib cage of the patient; another portion 189 is reflected. In
order for these back-scattered or reflected muscle wall waves to
add constructively at the feed point 171, the waves would have to
experience the same path lengths, in terms of integral multiples of
a wavelength, as for the paths of the waves scattered at the focal
point 172. For most of the unscattered waves that are reflected
from the breast-lung-rib cage interface, constructive addition at
the feed point 171 is quite unlikely. An arrangement as shown in
FIG. 10, therefore, suppresses unwanted returns or clutter from
muscles and from the patient's rib cage relative to the returns
that are scattered at the focal point of interest, point 172.
Other dielectric anomalies 190, such as might arise from a blood
vessel, will also scatter the incident millimeter wave power.
However, like the clutter returns from the muscle-rib cage, such
returns will be suppressed in amplitude or even omitted, relative
to the returns from the voxel containing the focal point 172.
Furthermore, since many ray paths are used, any minor and random
variations of the dielectric constant will tend to be averaged
out.
Other methods of discriminating the presence of a tumor from the
clutter scatter returns are possible. FIG. 11 illustrates one such
phenomenon, a resonant enhancement of the scattering cross section,
.sigma., that occurs when the circumference of a highly conductive
spherical scatterer equals the wavelength in the media around the
sphere. The cross-section relative to the projected area of the
sphere is shown as the ordinate 401. The abscissa 402 is the ratio
of the circumference to the wavelength. The curve 403 illustrates
how the cross section is enhanced by the resonant scattering that
takes place between the Rayliegh region 404 and the Mie (resonance)
region 405. In addition, internal resonances within the tumor are
possible. Despite the higher conductivity within the tumor, the
material within the tumor still behaves as a lossy dielectric
because of the very large value of its relative dielectric
constant. Therefore, internal resonances within the very high
dielectric constant tumor can be considered to occur where the
internal dimensions are in the order of a one half wave length--or
about 3 mm for an operating frequency of 10 GHz. Such resonances
can generate a unique response, quite different from those
generated from dielectric interfaces or other sources of clutter.
Such resonant responses can be observed by sweeping the frequency
over a wide bandwidth or exciting the breast tissues with a very
short duration mmw pulse and then observing the resonant
quasi-sinusoidal decay.
The foregoing description was aimed primarily at a prototype
suitable for clinical evaluations. A commercial version may avoid
the use of the boot and the elliptical reflector (FIG. 10). For
example, arrays of 6 mm rectangular waveguides may be filled with
dielectric material that has a relative dielectric constant similar
to that of the breast, roughly in the order of nine to sixteen. The
rectangular guide in the TE.sub.01 mode readily propagates 10 to 15
GHz frequencies. Each of the guides would be positioned in contact
with the breast, directly or through a very thin material used for
one of several standard brassieres. The phase angle of the power
presented to the guide-breast contact point would be identical to
the phase angle of each ray path, some of which paths are shown in
FIG. 10. For example, at positions 192 and 194 of FIG. 10, the
phase angle of the power at each of the waveguide exits would be
the same as the phase angle for each of ray paths 191 and 193
respectively. One hundred such 6 mm guides could be positioned in a
60 mm by 60 mm flat faced rectangular array to replace the
egg-shaped elliptical antenna 170 shown in FIG. 10. Given a
computer-aided ability to adjust the phase of the output power at
each of the guides, the position of each of the guides could be
made to fit the contours of many different breasts. The advantage
of this approach would be to permit mass screening, but at the
expense of a rather complex piece of equipment. The use of
computer-controlled functions and data analysis does make such an
approach feasible.
The foregoing can be better understood by referring to FIG. 13,
which shows a nine aperture wave guide module 450. Nine
double-ridged wave guides 451 are used. Each of these are filled
with a dielectric material 452 that approximates the relative
dielectric constant of normal breast tissue. In the case of a
screening system, only four wave guide apertures might be used. The
combination of modules pressed against the breast in place of the
dielectric plate 183 of FIG. 10. By proper phasing of the signals
to each of the wave guides, focal point can be positioned within
the breast without the need for mechanical movement.
FIG. 14 illustrates one way that the phase or timing of the signal
applied to the wave guides may be controlled to position the focal
point in a medium 418 which contains the aperture antennas 410A,
410B, 410C and 410D and focal points 412 and 413. A source 400 of
microwave power applies equiphased power via wave guides 401 and
402 to two power splitters 403 and 404. The outputs of the
splitters are applied, via wave guides 405A, 405B, 405C and 405D,
to the circulators or directional couplers 406A, 406B, 406C and
406D. The forward power through these devices is transferred via
the guides 407A, 407B, 407C and 407D to the variable time delay or
phase control devices 408A, 408B, 408C and 408D. The return power
is transferred via wave guides 416A, 416B, 416C and 416D to a
subsystem 417 that collects the returns in a format suitable for
additional processing by subsystem 255 of FIG. 6. The time delay in
each device 408 may be controlled by changing the magnetic field
bias applied to a ferrite element within each of the devices. Such
bias may be supplied via the cables 414A, 414B, 414C and 414D from
the time delay control subsystem 415. The outputs from wave guides
405 are controlled by the signal processing and display subsystem
255 of FIG. 6. Via wave guides 409A-409D, the time delayed or
phased controlled power is supplied to the aperture antennas
410A-410D. A portion of the outputs from these apertures reaches
the desired focal point 412 via pathways 411A, 411B, 411C and 411D.
At point 412, the phases of the rays shown are nearly
identical.
Assuming a time delay of t.sub.1, t.sub.2, etc. for each of the
delay control elements 408 and path lengths (411) d.sub.1, d.sub.2,
etc., then t.sub.1 +d.sub.1 /v=d.sub.4 /v for constructive addition
where v is the velocity of propagation in the medium 418. To meet
this requirement, t.sub.1 =(d.sub.4 -d.sub.1)/v. Other time delays
can be calculated in the same way.
Other methods of control are possible by controlling the phase of
the signals applied to each aperture instead of by the timing
devices. In this case, the relative phase between the signals
applied to apertures 411C and 411D can be redefined by noting the
following, where .omega. is the radian frequency [2 .pi.f] and
.theta..sub.12 is the phase difference between 411C and 411D, such
that .theta..sub.12 =.omega.[t.sub.2 -t.sub.1 ].
The confocal arrangement permits the scattered signals to return by
the same pathways as the applied wave form. These signals are
collected by the aperture antennas 410 and progress back through
the time delay devices 408 to the circulators 406. These, in turn
supply data on the scattered returns to subsystem 417.
FIG. 15 illustrates an alternate method of scanning the interior of
the breast. The microwave generation and signal recovery system 460
supplies power to an array of mechanically positionable wave guides
461A, 461B, 461C and 461D. Waveguides 461 are designed to slide
into guides 462 so that the distal end of guides 461 is in intimate
contact with the breast 463 on the chest 464 of an examination
subject. As noted before, the position of each guide can be
measured and this information can be used to calculate the timing
or phase data needed to position the focal point throughout the
breast. This method has the advantage that an interface plate such
as 183 of FIG. 10 is not needed to compress the breast 463, FIG. 15
and that better and more reproductible contact with the breast can
be made.
Dielectric materials in solid form are available with relative
dielectric constants that can exceed 100, that have relative low
losses, and that can be machined. These materials can be used to
fill the elliptical reflector or the waveguides (FIG. 10). Liquid
or slurry-like dielectrics with both low losses and dielectric
constants at 10 GHz in the order of ten may not be readily
available. However, some liquids, such as the silicones, have
dielectric constants of nearly three. Such oils could be mixed with
particles of materials that have dielectric constants that exceed
30 to 50 to form a slurry exhibiting a dielectric constant of the
order of nine. Conversely, acetone has a dielectric constant of 22
at ten GHz, and it could be mixed with a silicone oil to produce a
dielectric constant of nine for the mixture. Other possibilities
exist, including emulsions and similar techniques that allow
suspensions of one liquid in another or suspensions of particles in
a liquid.
The aforementioned techniques are not limited to backscatter; they
can be modified or augmented to detect both side scatter and
forward scatter. One forward scatter approach could use a
paddle-like source antenna and a paddle-like receiving antenna. At
least one of these would function similar to the antenna
illustrated in FIG. 10. For example, the more pendulous portion of
a breast can be placed between the paddles. This would permit
examination of a breast that is 100 mm thick with a system
optimized for a 50 mm penetration depth.
The above may be better understood by referring to FIG. 16. Here,
the breast 480 is positioned within two dielectric plates 472A and
472B. A cover plate 483 and gaskets 482, together with plates 472,
form a box-like structure that surrounds breast 480. The relative
dielectric constant of the box wall material is similar to that of
the breast. A thin plastic film 481 covers the portion of the
breast that is not in contact with the box. The space between this
plastic film and the breast is filled with a liquid that has the
same dielectric constant as the normal breast. A cable bundle 470
supplies microwave power to a series of waveguides 471 that are in
a housing 479A on plate 472A. Upon excitation, the power in these
guides is timed or phased such that the ray paths 474 come to a
focal point 476. The time delays in the guides 477 in the receiving
assembly 479B are timed such that any scattering occuring at point
476 will add constructively. The outputs of these guides are
carried to the signal processing subsystem via a cable bundle
471.
The aforementioned techniques may also be readily modified to
detect Changes in the plane of polarization. For example, a square
TE.sub.01 waveguide could inject a vertically polarized wave and
respond to a horizontally polarized wave. Similar arrangements
could be used for either side scatter or forward scatter
polarization anomaly sensing arrangements.
Another variation would be to use the illuminator and focusing
arrangements described above in combination with an "active" or
time domain method of separating the applied power from the
scattered power. Other such active or time domain methods utilize a
"chirp radar" to produce added resolution in depth and additional
clutter suppression. At a center frequency of 15 GHz a chirp radar
with a swept frequency bandwidth in the order of 5 GHz and with
phase correction for the dielectric behavior of the breast tissue
could produce range cell resolutions of the order of 10
millimeters. Alternatively, sequences of very short duration bursts
of 15 to 25 GHz waveforms should also provide isolation of the
applied power from the backscattered power by time gating
techniques. Burst durations in the order of 100 picoseconds will
provide depth discrimination of the order of 10 to 20 millimeters.
This added discrimination would not only suppress the incident
power, but also could suppress backscatter returns from the
different dielectric interfaces, such as the muscles around the rib
cage.
Active methods are of particular interest because these methods may
be functional with total path losses in excess of 100 dB. Such path
losses might be difficult to overcome with a passive system, since
it may be difficult to reduce clutter levels below 50 to 70 dB the
applied power. Since some of the clutter can be reduced by
considering only the returns in just one voxel, active systems
might be viable over a wider dynamic range. Also, shorter
wavelengths with greater resolution can be used, since active
systems can accept greater path losses, possibly as much as might
be experienced by a system with an operating frequency as high as
60 GHz.
To illustrate how time domain separation can be realized in broad
band pulse systems, FIG. 12 presents a further possible system 500.
Many of the components are similar to those noted in FIG. 6; they
are not repeated in FIG. 12. In system 500 the power and signal
direction functions of the isolator of FIG. 6 have been augmented
by a modulator 540 and a source 541 of 100 to 200 picosecond
pulses. In some systems, the isolator 224 may be omitted. A pulse
from the pulse source 541, via cable 543, gates on the modulator
540. This causes the modulator to generate a short burst of 15 GHz
sine waves that is applied, via a cable 242, to the input 225 of
the circulator 224. Also, the pulse source 541 supplies a timing
pulse to a blanker-modulator circuit 542 and to a signal processor
515. The blanker-modulator 542 suppresses any leakage of the
incident pulse through the isolator 224 from impinging on a
broad-band receiver 516. The timing pulse, via the cable 544, is
used by the signal processor 515 to determine the spatial position
of the different scattered returns by noting the time of arrival of
each of the returns. For example, the more distant returns that
might arise from the patient's rib cage would be delayed the most.
The combination of a pulsed sine wave source and a blanking
function (often called a transmit and receive function) essentially
provides a power and signal direction function that could replace
the circulator 224 function as illustrated in FIG. 6.
The pico-second-duration-pulse, time-domain system described for
FIG. 12 has some drawbacks that may be overcome by a
stepped-frequency, synthetic-time domain method. For example, the
noise level of the wide bandwidths needed to accommodate such short
duration pulses can be quite high. On the other hand, the
stepped-frequency method can have long well times at each
frequency, thereby reducing the bandwidth and noise level for the
signal processing system. While the confocal system is a powerful
tool to suppress the effect of some classes of heterogeneities, it
may not provide sufficient discrimination at deep penetration
depths. To mitigate this problem, a time gating technique can be
used to suppress scattered returns from shallow depths. Such a
method may note the presence of a weakly scattering tumor at depth.
If the relative dielectric constants of the intervening material
are uncertain, the geometrical position of the tumor cannot be
precisely determined. While this uncertainty poses a difficulty for
an imaging system, it should not affect the viability of a
screening system designed to detect abnormalities.
Swept frequency methods can be considered. For example, an FM Chirp
radar method that has been used in weapons detection systems
effectively separates desired returns from those generated by
system discontinuities. A version of this would be attractive in
conjunction with the confocal illumination method to separate the
effects of near surface discontinuities or hetrogeneities from the
returns at greater depth. Linear FM pulse compression radar (PCR)
techniques might also be considered. These have been described by
Jacobi (1986, reference seven hereafter) for biological imaging
applications. The theoretical resolution of a PCR is given by
.DELTA.R=C/2B, where C is the is the velocity of propagation in the
media, and B is bandwidth of the transmitted wave form. Assuming a
mid-band frequency of 8 GHz, a 5 GHz sweep and a medium with a
dielectric constant of nine, a range resolution of one cm is
indicated. However, a 2.5 GHz sweep may be more readily realized
and could produce an in-tissue resolution of two cm. To realize
this performance, the FM sweep must be highly linear, a pulse
compression filter developed for this application and the
dispersion effects of the dielectric compensated.
A stepped or swept frequency input impedance Fourier inversion
alternative exists. This option transforms data developed from the
frequency domain measurements to the time domain via digital
processing, thereby eliminating the need for a pulse compression
filter. This can be implemented by using either the confocal
illuminator of FIG. 10 or the phased array of FIG. 14. The output
signals from the circuit shown in FIG. 7 on lines 346 and 345 can
be viewed as a complex input impedance, S(j.omega.), at a radian
frequency of .omega.(.omega.=2 .pi.f) to the illuminator. As the
frequency is stepped from a low frequency to a higher frequency,
the complex input impedance for each frequency is stored in a
digital computer. If the frequency is swept or stepped over a band
similar to that noted for the PCR system, similar spatial
resolutions can be realized. Via digital processing, the complex
input impedance data is converted from the frequency domain to the
time domain using inverse Fourier transformation. The transformed
data is then in the form of an amplitude vs. time response, similar
to a radar A scope display, as if an impulse or stepped function
had been applied at port 234 of the circulator 224 in FIG. 7.
Initially, the returns from system discontinuities, such as from
connectors and the interface with the antenna in the illuminator,
will be displayed. Then, the reflections from anomalies in the
breast will be displayed, the reflections from the deeper anomalies
occurring at the longer times. The stepped frequency option offers
the opportunity to include a standard correction at each frequency
increment for a typical dispersion characteristic for normal breast
tissues and could also include compensation for other factors such
as path loss or system dispersion in the ferrite phase shifters.
Some of the more modern network analyzers include a built-in
stepped or swept frequency to time domain processing option.
The underlying mathematical basis is as follows. The general
Fourier transformations are: ##EQU1## Where F(f) is the impulse or
step response S(j.omega.) is the Fourier transformation of F(f)
.omega.=2 .pi. f, is time.
Throughout the foregoing specification and in the appended claims
the terms millimeter waves, or mm waves or mmw have been used to
generically represent the wavelengths of the electromagnetic waves
that propagate in the human breast tissue. Since the relative
dielectric constant of the breast is in the order of 9 to 12, the
free-space wave length will be reduced by a factor of three or
more. Thus, the in-tissue wavelengths over a frequency range of 3
to 60 GHz will range from about 30 mm to 1 mm.
As opposed to certain microwave hypothermia cancer treatment
technology, none of the technology presented here is intended to
heat significantly any portion of the breast. This requirement
limits the power deposition density onto the surface of the breast
to less than 10 milliwatts/cm.sup.2 and the volumetric heating rate
in any portion of the breast to less than 0.8 milliwatts per gram
of tissue as averaged over a time period of a few minutes. To
further assure minimal thermal effects, the input power is to be
turned off if the scanning system falters for any reason.
Other usages are as follows: The term impedance refers to the ratio
of the voltage to the current or of the electric field to the
magnetic field at a specified location. This term impedance is
qualified as "electrical" or "wave" respectively, depending on
whether voltages and currents or electromagnetic fields are
concerned. The term wave guide is used in the generic sense and
includes both cables and higher mode wave guides with just a single
transverse field. The terms effective aperture and effective focal
point are used in the generic sense wherein apertures and focal
points can be created physically or synthetically (such as often
used in synthetic aperture radar).
The effective focal point is not really a point but rather is
defined here as a region where the illuminating energy is most
concentrated in the breast. The effective focal point is further
defined as the region or volume where this energy concentration
occurs as affected by the heterogeneity of dielectric
characteristics of the normal breast tissues, the in-tissue
wavelength, the size and distance of the illuminating globular
aperture or the geometry and number of apertures used in a phased
array. The focal point positioning may be either mechanical or
electronic as in the case of a phased array.
The terms "detect" or "detection" are also used in the generic
sense, and may mean simply indicating the presence of a tumor or
more broadly providing data that permits imaging the location, size
and geometry of the tumor. Detecting, identifying, imaging or
locating a tumor also means noting the presence of an abnormality.
The terms "power and signal director" or "input power and signal
separation" are also used in a generic sense. Both passive and
active techniques not only enhance detection by suppressing the
direct effects of impinging power waves, but also can reduce false
signals or clutter. Such are introduced by imperfect matches
between impedances or by non-tumor scattering sources, such as the
breast/lung interface.
The following references are of utility in understanding the
foregoing specification:
Burdette, E. C., et. a1.(1980): In vivo measurement techniques for
determining dielectric properties at VHF through microwave
frequencies, IEEE Trans. on MTT, Vol MTT-28, No. 4 April, pp
414-427
Burdette, E. C., et. al. (1986): In situ permittivity at microwave
frequencies: perspective, techniques, results, medical applications
of microwave imaging, Medical Applications of Microwave Imaging,
Larsen, L. E. and J. H. Jacobi, IEEE press pp 13-40
Chaudhary, S. S., et. al. (1984): Dielectric properties of normal
and malignant human breast tissues at radiowave and microwave
frequencies, Indian Jr. of Biochemistry and biophysiscs, Vol. 21,
Feb pp76-79
Edrich, J., et. al. (1976): Complex permittivity and penetration
depth of muscle and fat tissues between 40 and 90 GHz, (1976) IEEE
Trans. MTT, vol. MTT-24, May pp273-275.
Johnson, E. C., et. al. (1972): Nonionizing electromagnetic wave
effects in biological materials and systems, Proc. of the IEEE,
Vol. 60, No. 6, June pp 694-695.
Kay, A. F. (1966): Millimeter wave antennas, Proc. of the IEEE,
Vol. 54, No. 4, pp 641-647
Larsen, E. L. and J. H. Jacobi, Eds. (1986): Medical Applications
of Microwave Imaging, IEEE press. Institute of Electrical and
Electronic Engineers, New York, pp. 138-147
Ramo, S., et. al. (1965): Fields and Waves in Communication
Electronics, John Wiley and Sons, New York
Rogers, J. A., et. al. (1983): The dielectric properties of normal
and tumor mouse tissue between 50 MHz and 10 GHz, British Jr. of
Radiology, vol. 56, May, pp 335-338.
Smith, W. J., (1966): Modern Optical Engineering, Mc Graw-Hill, New
York, N.Y.
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